Isolated DC-DC Voltage Converters

ABSTRACT

A switching voltage converter using an isolated topology includes a transformer for coupling power from an input source to an output load. The transformer must be protected to prevent saturation of its core due to excessive magnetic flux density as the transformer transfers power from its primary side to its secondary side. The magnetic flux is estimated using a voltage measured on the primary or secondary side of the transformer, wherein the secondary-side voltage may be a rectified voltage. If the estimated magnetic flux is detected as approaching a saturation level of the transformer core, any power being input to the transformer is curtailed. This may be accomplished by modifying pulse-width modulated (PWM) waveforms controlling power switches that control the input power transferred to the transformer. Using these techniques, transformer saturation may be avoided without requiring a significantly oversized transformer within the voltage converter.

TECHNICAL FIELD

The present application relates to isolated voltage converters and, in particular, relates to techniques for estimating and tracking the magnetic flux within a transformer of such a voltage converter, in order to prevent the transformer core from saturating.

BACKGROUND

Isolated direct-current (DC) to DC switching voltage converters use a transformer to convert power from an input source into power for an output load. Such voltage converters include primary-side power switches that convert DC input power into alternating current (AC) power that is fed to the primary side of a transformer. AC power supplied on the secondary side of the transformer is rectified to convert it back into DC power which, in turn, is provided to the output load. The primary-side power switches are typically controlled by pulse-width modulated (PWM) waveforms. A PWM controller generates the PWM waveforms with a frequency and duty cycle that are appropriate to meet the power needs of the output load.

The transformer in an isolated DC-DC voltage converter must be protected in order to prevent saturation of the transformer core and associated failure of the primary-side power switches. As the magnetic flux density within the transformer core approaches a saturation level, the external magnetic field can no longer efficiently increase the magnetization of the transformer core. The effect of this is that the primary winding of the transformer begins to appear as an electrical short circuit, which leads to excessive current through the primary winding. Such excessive current also flows through the primary-side power switches and can damage them. In order to avoid destroying the primary-side power switches and other problems that are associated with transformer core saturation, e.g., excessive heat, transformer core saturation must be prevented in DC-DC voltage converters.

The most direct technique for preventing core saturation is to measure the current flowing through the primary-side winding, and compare it against some current limit that indicates the core is saturating. If the primary-side current exceeds this limit, the PWM waveforms may be adjusted (e.g., a duty cycle of a PWM waveform may be reduced) to prevent the core from saturating. This technique requires sensing the primary-side current, which requires additional circuitry and which typically has some associated power loss. While such a technique is effective and may also be used to balance the half cycles of current and flux, it may not be feasible in some applications. In particular, this technique is not appropriate in isolated DC-DC voltage converters wherein the PWM generator and/or controller is located on the secondary side of the transformer.

Without active prevention of core saturation, as described above, a transformer core is susceptible to flux walkaway, in which small mismatches in the positive and negative half cycles of the voltage converter lead to a gradual increase in the flux magnitude which, eventually, leads to saturation of the transformer core. This can be addressed by balancing the positive and negative half cycles. One technique for doing so is to couple power into the primary-side winding using capacitors. This is often not a preferred technique, due to the added circuitry (size), component cost, power loss, etc., as well as that such a technique does guarantee safe operation. Other flux-balancing techniques, which may operate in conjunction with or as alternatives to capacitor usage, serve to balance positive and negative half cycles over a fairly large time scale, but do not immediately recognize and prevent core saturation. Because such flux-balancing techniques are fairly slow acting, the average transformer flux will tend to rise to positive values or fall to negative values, before the flux-balancing techniques are able to compensate for such excursions. In order to ensure a transformer core does not saturate when using such slow-acting flux balancing, the transformer must be designed with a significantly higher flux saturation level than would be required if perfect flux balancing were available. This may be done by choosing a transformer having an air gap or that is physically larger (e.g., having a larger core cross-sectional area) than otherwise necessary, in order to achieve an adequate safety margin for the flux saturation. Such an overdesigned transformer should be avoided in most applications, due to, e.g., its increased size and increased cost.

Accordingly, there is a need for improved techniques for estimating magnetic flux within the transformer of a DC-DC voltage converter, for immediately preventing saturation of the transformer core, and for balancing the positive and negative flux excursions within the transformer. Such techniques should be feasible for implementation on the primary or the secondary side of the voltage converter, and should not require sensing the primary-side current. Use of such techniques should allow isolated DC-DC voltage converters to be designed with smaller and more efficient transformers, while achieving safe operation that avoids transformer core saturation.

SUMMARY

According to an embodiment of a switching voltage converter, the voltage converter includes a power stage, a transformer, a conditioning circuit, and a controller. The power stage is coupled to an input power source and includes one or more power switches. The transformer includes primary and secondary windings, with the primary winding coupled to the power stage. The conditioning circuit couples the secondary windings of the transformer to an output node that is operable to supply power to a load of the voltage converter. The controller is operable to generate pulse-width modulated (PWM) waveforms for controlling the power switches of the power stage, wherein each PWM waveform is comprised of a series of PWM pulses. The controller is also operable to estimate the magnetic flux within the transformer based upon a voltage within the voltage converter. This voltage may be taken across the primary winding of the transformer, across the secondary winding of the transformer, or elsewhere within the conditioning circuit. The estimated magnetic flux is used to detect an overflux condition in which the estimated magnetic flux has exceeded a flux magnitude limit for the transformer. If such a condition is detected, a pulse within the PWM waveforms is truncated before the PWM waveforms are provided to the one or more power switches.

According to a method within a voltage converter, magnetic flux saturation within the core of a transformer is avoided by estimating the transformer's magnetic flux and curtailing power input to the transformer if the estimated magnetic flux approaches a saturation limit. The method includes the step of generating pulse-width modulated (PWM) waveforms for controlling one or more power switches within the voltage converter, wherein each PWM waveform is comprised of a series of PWM pulses. The magnetic flux of the transformer is estimated based upon a voltage across the primary winding of the transformer, a voltage across the secondary winding of the transformer, or a voltage elsewhere on the secondary side of the voltage converter. If the estimated magnetic flux exceeds a flux magnitude limit for the transformer, an overflux condition is detected. In response to detecting such an overflux condition, one or more pulses within the generated PWM waveforms are truncated in order to temporarily disable power from being input to the transformer core. The modified PWM waveforms are provided to the power switches.

Those skilled in the art will recognize additional features and advantages upon reading the following detailed description, and upon viewing the accompanying drawings.

BRIEF DESCRIPTION OF THE FIGURES

The elements of the drawings are not necessarily to scale relative to each other. Like reference numerals designate corresponding similar parts. The features of the various illustrated embodiments can be combined unless they exclude each other. Embodiments are depicted in the drawings and are detailed in the description that follows.

FIG. 1 illustrates a circuit diagram of a voltage converter using a full-bridge topology, wherein the voltage converter is configured to estimate magnetic flux within a transformer and to modify PWM waveforms to prevent saturation of the transformer core.

FIG. 2 illustrates waveforms corresponding to PWM control signals, actual magnetic flux, and estimated magnetic flux within a voltage converter such as that shown in FIG. 1.

FIG. 3 illustrates waveforms similar to those of FIG. 2, but also illustrates detection of a high-flux condition and the resultant modification of the PWM waveforms.

FIG. 4 illustrates waveforms corresponding to a transformer input voltage, the actual magnetic flux of the transformer, and an estimated magnetic flux of the transformer, for a situation in which the input to the transformer includes a step increase in its voltage.

FIG. 5 illustrates a circuit diagram for a voltage converter similar to that of FIG. 1, except that the flux estimation within the voltage converter of FIG. 5 is based upon a voltage across the secondary windings of the transformer.

FIG. 6 illustrates a circuit diagram for a voltage converter similar to that of FIG. 5, except that the flux estimation within the voltage converter of FIG. 6 is based upon a rectified voltage on the secondary side of the voltage converter.

FIG. 7 illustrates waveforms for a transformer input voltage, actual magnetic flux of the transformer, a secondary-side rectified voltage, and a flux estimate based upon the rectified voltage, wherein the waveforms correspond to waveforms that may be found within the voltage converter of FIG. 6.

FIG. 8 illustrates waveforms similar to those of FIG. 7, but also illustrates a situation in which the input to the transformer includes a step increase in its voltage.

FIG. 9 illustrates a more detailed version of a flux controller and a PWM generator, as are included in the voltage converters of FIGS. 1, 5, and 6.

FIG. 10 illustrates a flux controller and PWM generator similar to those of FIG. 9, but also including a fast duty cycle adjustment.

FIG. 11 illustrates PWM waveforms similar to those of FIG. 3, except that the waveforms are phase shifted to control the amount of power transfer, rather than using duty cycles to control the amount of power transfer.

FIG. 12 illustrates a voltage converter using an active clamp forward (ACF) topology, and which uses flux estimation and overflux prevention techniques as described for the full-bridge voltage converters.

FIG. 13 illustrates a method within a voltage converter for estimating flux within a transformer of the voltage converter and for avoiding flux saturation within the transformer.

DETAILED DESCRIPTION

The embodiments described herein provide techniques for estimating magnetic flux within a transformer core of an isolated DC-DC voltage converter. The estimated magnetic flux is continually tracked and, if it approaches a flux saturation limit of the transformer, a controller of the voltage converter immediately curtails the power being input to the transformer. This may be accomplished, e.g., by modifying pulse-width modulated (PWM) waveforms that control power switches that provide current to a primary winding of the transformer. The PWM waveforms may be modified with very little delay meaning that it is not necessary to have a large safety margin in order to prevent transformer core flux saturation. This, in turn, means that a smaller transformer may be used as compared with DC-DC voltage converters that do not use such flux estimation and tracking techniques.

The flux estimation described herein may also be used for flux balancing, e.g., in a slow control loop. While the flux estimation, flux tracking, and flux limiting techniques described herein make flux balancing less important, at least for preventing core saturation, it is still desirable to maintain an average flux density near zero. The average magnetic flux could drift to non-zero values due to implementation issues such as timing mismatches between the positive and negative half cycles, a change in the load requirements, or a DC offset for the average voltage applied to a primary-side winding of the transformer. By maintaining a running average of the flux estimation, a long-term non-zero average flux may be identified, and the controller can adapt the PWM waveforms to drive this long-term average flux to zero.

The flux estimation techniques described below do not rely upon sensing a current on the primary-side of an isolated DC-DC voltage converter. Instead, the flux is estimated using voltages sensed at various nodes within the DC-DC voltage converter. More particularly, the techniques described below estimate flux using a voltage corresponding to the transformer's primary winding, a voltage corresponding to the transformer's secondary winding, or a rectified voltage on the secondary-side of the DC-DC voltage converter.

The flux estimation and tracking is performed within a controller of the DC-DC voltage converter. This controller also includes a PWM generator, which provides the signals used to control the power switches on a primary side of the DC-DC voltage converter. If the controller detects that the flux estimation is nearing a flux saturation limit, the controller will modify the PWM signals to curtail further power from being input to the transformer and, thereby, prevent the transformer core from reaching a saturation point. The techniques presented herein are particularly appropriate for a controller located on the secondary side of a DC-DC voltage converter, but could be readily extrapolated to a controller implemented on the primary side of such a converter.

The techniques described herein are not limited to single-phase or multi-phase voltage converters. For clarity in the following description, the techniques are described in the context of a single-phase voltage converter, but it should be appreciated that the techniques are readily extrapolated to multi-phase voltage converters. Furthermore, the techniques apply to both fixed and variable-frequency DC-DC voltage converters. For clarity in the following description, voltage converters using a fixed switching frequency are shown, but it should be appreciated that the techniques could be applied to variable-frequency voltage converters.

Various embodiments of voltage converter circuits and methods within voltage converters are provided in the following detailed description and the associated figures. The described embodiments provide particular examples for purposes of explanation, and are not meant to be limiting. Features and aspects from the example embodiments may be combined or re-arranged, except where the context does not allow this.

Three exemplary embodiments of voltage converter circuits are described in the following. These embodiments vary primarily in the techniques used for estimating the magnetic flux of a transformer within a DC-DC voltage converter. In a first of these embodiments, the voltage across a primary winding of the transformer is used for estimating the magnetic flux. In a second embodiment, the voltage across a secondary winding of the transformer is used for estimating the magnetic flux. In a third embodiment, a rectified voltage on the secondary side of the transformer is used for estimating the magnetic flux. These embodiments are described for voltage converters using a full-bridge topology, but the techniques are also applicable to other topologies. A variation of the third embodiment is described to show how the techniques may be used within an active clamp forward topology. In addition to the voltage converter embodiments, an embodiment of a method within a voltage converter is also described.

FIG. 1 illustrates a DC-DC voltage converter 100 within which magnetic flux estimating, limiting, and balancing techniques may be implemented. The illustrated voltage converter 100 is a full-bridge converter, but the techniques also apply to other push-pull topologies, active clamp forward topologies, etc. The voltage converter 100 includes a power stage 110, a transformer 120, an isolator 130, a conditioning circuit 140 and a controller 160. An input power source V_(IN) provides power to the voltage converter 100, and the voltage converter 100 supplies output power to a load 150.

The input power source V_(IN) is provided to the power stage 110, which couples it to the transformer 120 using power switches. The power stage 110 includes four power switches Q₁, Q₂, Q₃, Q₄, each of which has an associated driver within a driver stage 112. The switches Q₁, Q₂, Q₃, Q₄ are oriented in a full-bridge configuration. During an active interval within a positive half-cycle of the voltage converter 100, switches Q₁ and Q₃ are conducting, thereby producing a positive voltage across V_(AB) that is provided to the transformer 120. During an active interval within a negative half-cycle of the voltage converter 100, switches Q₂ and Q₄ are conducting, thereby providing a negative voltage to the transformer 120 across its input V_(AB). Additionally, there may be “dead time” intervals during which none of the switches Q₁, Q₂, Q₃, Q₄ are conducting and no voltage is provided to the transformer 120 across V_(AB).

The power switches Q₁, Q₂, Q₃, Q₄ are illustrated in FIG. 1 as enhancement-mode metal-oxide semiconductor field-effect transistors (MOSFETs), but other switch types may be used. For example, junction field-effect transistors (JFETs), bipolar junction transistors (BJTs), insulated gate bipolar transistors (IGBTs), high electron mobility transistors (HEMTs), or other types of power transistors may be preferred in some applications. The power switches Q₁, Q₂, Q₃, Q₄ may be integrated on the same semiconductor die, may each be provided on separate dies, or may otherwise be spread across a plurality of semiconductor dies. The drivers within the driver stage 112 may be integrated on the same semiconductor die(s) as their corresponding switches Q₁, Q₂, Q₃, Q₄, or may be provided on separate dies.

The transformer 120 includes a primary winding 122 having N1 turns, secondary windings 124 a, 124 b having N2 turns each, and a core 126. The transformer 120 of FIG. 1 also includes a leakage inductance L_(LK), which is not a separate component but which models stray inductance that is not included in the windings 122, 124 a, 124 b. The secondary windings 124 a, 124 b are connected together at a center tap. A rectified voltage node V_(rect) is coupled to this center tap. Presuming the effect of the leakage inductance L_(LK) to be insignificant, the ratio N2/N1 determines the ratio of the rectified voltage V_(rect) to the input voltage V_(AB) of the transformer 120.

The conditioning circuit 140 is configured to rectify the voltage output from the secondary windings 124 a, 124 b and to filter the rectified voltage V_(rect) before it is provided to the load 150. As shown in FIG. 1, rectification switches Q_(SR1), Q_(SR2) are controlled by the controller 160 to produce the rectified voltage V_(rect) from the AC voltage induced across the secondary windings 124 a, 124 b. (The rectified voltage V_(rect) may need to be shifted, e.g., using a resistor divider, before being input to the controller 160. For ease of illustration, this is not shown.) Other rectification circuits or techniques may be used. For example, diodes may couple each outer terminal of the secondary windings 124 a, 124 b to a rectified voltage node, while the center tap is coupled to a ground of the load 150. In another alternate configuration, four diodes in a bridge configuration may be used with a secondary winding that has no center tap. In general, such diode-based rectification is not preferred for low voltages due to the power loss associated with the diodes, as compared with the active rectification using power switches Q_(SR1), Q_(SR2) as shown in FIG. 1. The conditioning circuit 140 also includes an output inductor L_(O) and capacitor C_(O) which form an LC filter. The LC filter serves to smooth the voltage V_(O) provided to the load 150.

The controller 160 is responsible for controlling the voltage converter 100 in order to supply the necessary power (voltage V_(O) and current I_(LOAD)) to the load 150. This includes controlling the rectification switches Q_(SR1), Q_(SR2) to generate the rectified voltage V_(rect), and generating PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q4) that control the switches Q₁, Q₂, Q₃, Q₄ of the power stage 110. Techniques for controlling rectification switches are well-known in the art, and such conventional techniques are not described here in order to avoid obscuring the unique aspects of this invention. The PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q4) that control the power switches Q₁, Q₂, Q₃, Q₄ are generated to ensure the load 150 is supplied adequate power, and this generation is typically based upon the output voltage V_(O) and/or the load current I_(LOAD). Conventional techniques are used to generate baseline PWM waveforms, based upon load requirements. For example, a proportional, integral and derivative (PID) controller might use the output voltage V_(O) to adaptively determine duty cycles for the PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q4). Because such techniques are well-known, they will not be described further herein. (The output voltage V_(O) may need to be shifted, e.g., using a resistor divider, before being input to the controller 160. For ease of illustration, this is not shown.) Instead, the following description focuses on the unique aspects of this invention, which are directed to techniques for modifying the PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q4) in order to prevent saturation of the transformer core 126, wherein the PWM waveform modification is based upon an estimation of flux within the transformer core 126.

The controller 160 and its constituent parts may be implemented using a combination of analog hardware components (such as transistors, amplifiers, diodes, and resistors), and processor circuitry that includes primarily digital components. The processor circuitry may include one or more of a digital signal processor (DSP), a general-purpose processor, and an application-specific integrated circuit (ASIC). The controller 160 may also include memory, e.g., non-volatile memory such as flash, that includes instructions or data for use by the processor circuitry, and one or more timers. The controller 160 inputs sensor signals such as signals corresponding to V_(O), V_(rect), and I_(SENSE).

The voltage converter controller 160 includes a flux controller 170 and a PWM generator 180. The flux controller 170 is configured to estimate and track the magnetic flux of the transformer 120, to limit this magnetic flux by altering the PWM waveforms V_(PWMN) _(_) _(Q1), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q4) generated by the PWM generator 180, and, optionally, to balance the magnetic flux by driving its long-term average to zero. These techniques are initially described using the waveforms of FIGS. 2, 3, and 4. More detailed descriptions of an exemplary flux controller and an exemplary PWM generator are provided in FIGS. 9 and 10.

The change in the magnetic flux density (B) within a transformer core over a time interval T_(x) is given by:

$\begin{matrix} {{{\Delta \; B} = \frac{\int_{t_{0}}^{t_{0} + T_{x}}{{v(t)}\ {dt}}}{NA}},} & (1) \end{matrix}$

where v(t) is the voltage across a winding of the transformer,

N is the number of turns of the transformer winding, and

A is the cross-sectional area of the transformer.

Assuming to is the beginning of a switching cycle of the voltage converter 100, and T_(x) is the switching period (i.e., the inverse of the switching frequency), the flux density change over the period T_(x) is ideally zero. This occurs when the positive flux excursion occurring during a positive half-cycle of the voltage converter is perfectly balanced with the negative flux excursion occurring during a negative half-cycle of the voltage converter. Such perfect balance between the positive and negative excursions may be disrupted for various reasons including, e.g., a load release that decreases the PWM duty cycle, a load step that increases the PWM duty cycle, and a change in the source voltage V_(IN) that is coupled to the transformer 120.

Considering the primary side of the transformer 120 and assuming the leakage inductance L_(LK) is insignificant, the flux change of equation (1) may be rewritten as:

ΔBN ₁ A=∫ _(t) ₀ ^(t) ⁰ ^(+T) ^(x) ν_(AB)(t)dt,  (2)

where N₁ is the number of turns in the primary winding 122,

A is the cross-sectional area of the transformer 120, and

V_(AB)(t) is the voltage across the primary side of the transformer 120.

Converting equation (2) into discrete time wherein the voltage V_(AB) is sampled using a sample clock having a period T leads to:

ΔBN ₁ A=T*Σ _(k) ₀ ^(k) ⁰ _(+K)ν_(AB)(k), over the period from k ₀ to k ₀ +K.  (3)

The right-hand sides of equations (2) and (3) may be considered to provide variants of the magnetic flux change, wherein the variants are provided in Volt-seconds. Design parameters for the number of turns N₁ of the primary winding 122, the effective core area A of the transformer 120, and the flux density saturation limit BSAT are stored in the controller 160. For example, the controller 160 may contain a non-volatile memory (not shown) for storing these values, and the values may be loaded into the memory during a configuration or calibration stage of the voltage converter 100. Given these parameters, an upper saturation limit given by B_(SAT)N₁A and a lower saturation limit given by −B_(SAT)N₁A, both of which are in Volt-seconds, may be used to indicate an overflux condition of the transformer core 126.

FIG. 2 illustrates the magnetic flux B in the transformer core 126 over three cycles of the voltage converter 100, as well as an estimation of the magnetic flux as tracked in the controller 160. These waveforms 200 illustrate operation during which the magnetic flux B is confined within saturation limits B_(SAT) _(_) _(HI), B_(SAT) _(_) _(LO) (B_(SAT) _(_) _(HI)=B_(SAT), B_(SAT) _(_) _(LO)=−B_(SAT)). In a sub-embodiment of a voltage converter corresponding to the illustrated waveforms 200, a counter within the flux controller 170 is used to estimate the magnetic flux B. Whenever the primary-side voltage V_(AB) is detected as being high (positive), the counter is incremented, whereas the counter is decremented whenever the primary-side voltage V_(AB) is detected as being low (negative). The counter is unchanged if the primary-side voltage V_(AB) is at or near zero. The determination of whether the primary-side voltage V_(AB) is high, low or near zero is performed by the flux controller 170, which, as shown in FIG. 1, inputs voltages corresponding to nodes A and B via the isolator 130. In this sub-embodiment, the implementation of equation (3) is effectively simplified to assume a constant value for V_(IN), and that the magnitude of V_(AB) is equivalent to this constant value, as indicated in the following variation of equation (3):

$\begin{matrix} {{{\Delta \; {BN}_{1}A} = {v_{I\; N}T*{\sum\limits_{k_{0}}^{k_{0} + K}{\delta_{{AB}\;}(k)}}}},{{{wherein}\mspace{14mu} {\delta_{AB}(k)}} = \left\{ {\begin{matrix} {1,} & {{{if}\mspace{14mu} {v_{AB}(k)}} > v_{AB\_ THRESH}} \\ {{- 1},} & {{{if}\mspace{14mu} {v_{AB}(k)}} < {- v_{{AB\_ THRESH}\;}}} \\ {0,} & {otherwise} \end{matrix}.} \right.}} & (4) \end{matrix}$

In equation (4), the threshold V_(AB) _(_) _(THRESH) is chosen to be at some value between 0 and an expected value of V_(IN), e.g., V_(AB) _(_) _(THRESH) could be

$\frac{v_{IN}}{2}.$

The PWM generator 180 provides PWM waveforms 210, 220 that control the power switches Q₁, Q₂, Q₃, Q₄. During a positive interval of each cycle, a PWM pulse is generated on the control signals V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q3) in order to enable the power switches Q₁ and Q₃, as exemplified by the pulse 212 during cycle 1. During a negative interval of each cycle, a PWM pulse is generated on the control signals V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q4), in order to enable the power switches Q₂ and Q₄, as exemplified by the pulse 224 during cycle 1. This leads to positive and negative voltage pulses across V_(AB), such as the pulses 232, 234 during cycle 1. Due to circuit delays through the isolator 130, the driver stage 112, and the power switches Q₁, Q₂, Q₃, Q₄, the voltage pulses across V_(AB) are slightly delayed relative to the PWM control signals V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q4) output by the PWM generator 180.

The magnetic flux B changes over time as illustrated in the waveform 240. A first increase 242 in the flux is generated by the first positive voltage pulse 232 across V_(AB). This is followed by a first flux decrease 244 that corresponds to the first negative voltage pulse 234 across VA. The duty cycles of the PWM waveforms 210, 220, increase during cycles 2 and 3 due, e.g., to an increased power requirement of the load 150. As illustrated, an (undesirable) positive bias develops for the magnetic flux B during cycles 2 and 3.

A counter located in the flux controller 170 increments whenever the voltage V_(AB) is detected as being positive, and decrements whenever the voltage V_(AB) is detected as being negative. The counter effectively tracks a variant of the value described in equation (4). A waveform 250 corresponding to the resultant count is illustrated in FIG. 2, and it can be seen that this Count estimates the actual magnetic flux B waveform 240. Count limits Count_(LIM) _(_) _(HI), Count_(LIM) _(_) _(LO) corresponding to the magnetic flux limits B_(SAT) _(_) _(HI), B_(SAT) _(_) _(LO) are also shown in the Count waveform 250. The count limits may be given by:

$\begin{matrix} {{{Count}_{LIM\_ HI} = {\frac{N_{1}*A*B_{SAT\_ HI}}{T*v_{IN}} - \Delta}},{{Count}_{LIM\_ LO} = {\frac{N_{1}*A*B_{SAT\_ LO}}{T*v_{IN}} + {\Delta.}}}} & (5) \end{matrix}$

The flux limits B_(SAT) _(_) _(HI), B_(SAT) _(_) _(LO) may be set to, e.g., a saturation flux level +/− BSAT of the transformer core 126 and the increment Δ represents a safety margin to ensure the magnetic flux limits B_(SAT) _(_) _(HI), B_(SAT) _(_) _(LO) are not actually reached due to practical considerations such as, e.g., circuit delays.

The waveforms 200 illustrated in FIG. 2 show how a counter may be used to estimate the magnetic flux, but do not address any actions taken if the magnetic flux magnitude, or an estimate thereof, exceeds some threshold. Such a situation is illustrated in the waveforms 300 of FIG. 3. These waveforms 300 are similar to the waveforms 200 of FIG. 2, except that the counter, which estimates the magnetic flux B, reaches a count limit and, as a result, the PWM waveform 310 is modified to curtail the power input to the transformer 120.

At time t=t_(EXC), the Count reaches or exceeds the upper count limit Count_(LIM) _(_) _(HI). This is detected by the flux controller 170 which, in response to said detection, indicates to the PWM generator 180 that it should promptly curtail any power being input to the transformer 120. In response to this indication, the PWM generator 180 clamps the ongoing positive pulse 313 within cycle 3. Stated alternatively, the pulse 313 is shortened (truncated) relative to what it would have been without detecting a high-flux condition. Note that there is a slight delay between the detection at time t=t_(EXC) and the falling edge of the pulse 313. Shortly after the falling edge of PWM pulse 313, the power switches Q₁ and Q₃ are disabled, and the input source voltage V_(IN) is disconnected from the transformer input voltage V_(AB), as indicated by the falling edge of the positive V_(AB) pulse 335 within cycle 3. At this point, the magnetic flux B stops rising, as does the magnetic flux estimation tracked by the Count waveform 350. Note that while the count limit Count_(LIM) _(_) _(HI) is briefly exceeded, the magnetic flux B stays below the flux limit B_(SAT) _(_) _(HI). The negative pulse 337 of the V_(AB) waveform during cycle 3 is unaffected by any clamping. Over the 3 cycles illustrated in FIG. 3, the magnetic flux waveform 340 and the Count waveform 350 exhibit a positive bias (average), but the clamping serves to reduce this bias relative to an embodiment in which there is no clamping.

As described thus far, the flux controller 170 uses a counter with a fixed increment/decrement to estimate the magnetic flux B. While such an implementation may work well when the input voltage V_(IN) is very stable, problems may occur if there is variation in the input voltage V_(IN). Such a situation is illustrated in the waveforms 400 of FIG. 4. For ease of illustration, the PWM control signals V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q3). V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q4) are not shown, but it should be understood that these control signals are as explained above in FIG. 2 and FIG. 3.

Whereas FIGS. 2 and 3 illustrate a situation wherein an increase in the power required by the load 150 (i.e., a load step) causes increasing V_(AB) pulse intervals, the V_(AB) pulse intervals of FIG. 4 are relatively stable. However, a step change 431 in the magnitude of the V_(AB) pulses occurs during cycle 2. Such a step change 431 may occur due to an increase in the source voltage V_(IN). Responsive to the increased magnitude 431 of the V_(AB) pulses, the rate of change (slope) of the magnetic flux B increases 441. If the counter used for estimating this flux uses a fixed increment/decrement, as in the sub-embodiment corresponding to the waveforms of FIG. 3, the resultant count will not account for the increased voltage V_(IN), the corresponding increase in the V_(AB) pulse magnitudes, and the resultant magnetic flux B increase. In turn, the flux estimation provided by the counter will not accurately track the actual magnetic flux B meaning that either the flux limits B_(SAT) _(_) _(HI), B_(SAT) _(_) _(LO) may be exceeded or that a large safety margin, e.g., a large value for the Δ parameter mentioned in the prior sub-embodiment, is required when determining the count limits Count_(LIM) _(_) _(HI), Count_(LIM) _(_) _(LO).

In a further sub-embodiment, the above problems are addressed by using a variable increment/decrement for the counter, which provides a more accurate flux estimate and which accounts for variation in the input source voltage V_(IN). Such an embodiment more closely implements the flux estimation of equation (3), as opposed to the simplified implementation associated with equation (4). The improved flux estimate (Count) is given by:

Count=ΔBN ₁ A=T*Σ _(k) ₀ ^(k) ⁰ ^(+K)ν_(AB)(k), over the period from k ₀ to k ₀ +K.  (6)

The waveforms 400 resulting from a sub-embodiment making use of such an improved flux estimate are shown in FIG. 4. Note that the count limits Count_(LIM) _(_) _(LO), Count_(LIM) _(_) _(HI) are modified such that they are no longer normalized by an expected input voltage V_(IN). Hence, these limits may be given by:

$\begin{matrix} {{{Count}_{LIM\_ HI} = {\frac{N_{1}*A*B_{SAT\_ HI}}{T} - \Delta}},{{Count}_{LIM\_ LO} = {\frac{N_{1}*A*B_{SAT\_ LO}}{T} + {\Delta.}}}} & (7) \end{matrix}$

According to the waveform 430 illustrated in FIG. 4, the voltage V_(AB) provided to the transformer 120 has a step increase 431 in its value during a positive interval of cycle 2. This causes an increase in the rate 441 at which the magnetic flux B is increasing, as shown in the flux waveform 440. The flux estimation based upon a Count as given by equation (6) tracks 451 this increased magnetic flux rate 441. The Count waveform 450 does not reach the upper count limit Count_(LIM) _(_) _(HI) during cycle 2. However, the increased magnitude of the voltage V_(AB) causes the improved count to drop below the lower count limit Count_(LIM) _(_) _(LO) at time t=t_(EXC) during the negative interval of cycle 2. As in the sub-embodiment described in relation to FIG. 3, detection that the flux estimation (Count) reaches a count limit Count_(LIM) _(_) _(LO), Count_(LIM) _(_) _(HI) causes the flux controller 170 to provide an indication to the PWM generator 180 that any ongoing PWM pulse should be clamped. This results in the negative VA pulse 433 during cycle 2 being shortened relative to the PWM pulse that would be generated if no high-flux condition were detected. While the flux estimation given by Count falls below the lower limit Count_(LIM) _(_) _(LO), the magnetic flux B of the transformer core 126 stays bounded within the flux limits B_(SAT) _(_) _(HI), B_(SAT) _(_) _(LO).

The above sub-embodiments describe that a Count used to estimate magnetic flux B may use a fixed increment/decrement or may use an increment/decrement determined by a voltage V_(AB) sampled on each clock period of the Count. In yet another sub-embodiment, the increment/decrement may be based upon the voltage V_(AB) (or the associated input voltage V_(IN)), but it may be sampled at a rate less than that of the clock used for the Count. For example, the voltage V_(AB) (or the input voltage V_(IN)) may be sampled once per switching cycle, and the resultant voltage used by the counter for the next switching cycle. In a variant of this sub-embodiment, the voltage across V_(AB) during positive and negative half cycles may be integrated or averaged, and the results used as the increment/decrement amount for the next switching cycle of the voltage converter.

FIG. 5 illustrates a second embodiment of a voltage converter 500. Whereas the above sub-embodiments are based upon a first embodiment in which the magnetic flux B is estimated using the voltage V_(AB) across the input to the transformer 120, the embodiment of FIG. 5 uses the voltage V_(CD) across the secondary windings 124 a, 124 b of the transformer 120. The voltage converter 500 of FIG. 5 is similar to the voltage converter 100 of FIG. 1, and only those components that are significantly different are described below.

Because the flux estimation techniques of the voltage converter 500 do not use the voltage V_(AB) corresponding to the transformer 120 input, the isolator 530 is simplified as it need not transfer voltages corresponding to nodes A and B from the primary to the secondary sides of the voltage converter 500. Voltages corresponding to nodes C and D are provided to a flux controller 570 within a controller 560. These voltages V_(C), V_(D) may be sensed within the conditioning circuit 540, within the transformer 120, or somewhere in between. The controller 560 and the flux controller 570 therein are largely the same as the corresponding circuits 160, 170 within the voltage converter 100 of the first embodiment, except as explained below.

The magnetic flux change for the transformer core 126 may be given by:

ΔBN ₂ A=∫ _(t) ₀ ^(t) ⁰ ^(+T) ^(x) ν_(CD)(t)dt,  (8)

-   -   where N₂ is the number of turns in one of the secondary windings         124 a, 124 b,     -   A is the cross-sectional area of the transformer 120, and     -   V_(CD)(t) is the voltage across the secondary windings 124 a,         124 b of the transformer 120.         Note that equation (8) represents a variation of equation (2),         the variation being that the magnetic flux change AB is based         upon parameters for the secondary side of the transformer 120         rather than on its primary side. Equation (8) can be converted         into discrete time wherein the voltage V_(CD) is sampled using a         sample clock having a period T, thereby leading to:

ΔBN ₂ A=T*Σ _(k) ₀ ^(k) ⁰ ^(+K)ν_(CD)(k), over the period from k ₀ to k ₀ +K.  (9)

Sub-embodiments that estimate magnetic flux B based upon equation (9) may be implemented in a manner similar to the sub-embodiments described in conjunction with the voltage converter 100 of FIG. 1. For example, a sub-embodiment may use a counter that increments/decrements by a fixed amount, as described previously regarding FIG. 2, FIG. 3, and equation (4). Another sub-embodiment may use a counter that increments/decrements by a value corresponding to the secondary-side voltage V_(CD), in a manner analogous to that described in relation to FIG. 4 and equation (6). Due to their similarities with the sub-embodiments of the first embodiment, these sub-embodiments of the second embodiment are not described in detail here. The techniques of the second embodiment are the same as those of the first embodiment except that the flux estimation, as implemented within the flux controller 570, is based upon the secondary-side voltage V_(CD) and the turns N₂ of the secondary windings 124 a, 124 b. Note, also, that the count limits Count_(LIM) _(_) _(HI), Count_(LIM) _(_) _(LO), e.g., as given by equations (5) and (7), are altered to use the secondary-side parameters V_(CD), N₂ The safety margin given by Δ may also need to be altered to account for, e.g., smaller voltages on the secondary side of the voltage converter 500 as compared to the primary side (for a step-down converter), and/or the differing delays in sensing the voltage across V_(CD) as compared to V_(AB).

FIG. 6 illustrates a voltage converter 600 according to a third embodiment. This third embodiment uses voltages on the secondary side of the voltage converter 600 for estimating the magnetic flux within the transformer core 126. However, the voltage converter 600 of this embodiment uses a rectified voltage, such as V_(rect), rather than a (signed) voltage V_(CD) across the secondary winding, in estimating the magnetic flux B. This third embodiment is considered preferred since it does not require sensing additional voltages such as V_(AB) or V_(CD). As illustrated in FIG. 6, the rectified voltage V_(rect) is already input to the controller 660 for purposes of voltage rectification. This voltage V_(rect), may also be provided to the flux controller 670 where it can be used for flux estimation.

The rectified voltage V_(rect), does not inherently indicate the polarity of the magnetic flux B within the transformer core 126. While the flux polarity could be found by sensing winding voltages V_(AB) or V_(CD), the polarity can more easily be obtained from the PWM generator 680. For example, the flux polarity B_(POL) may be considered positive whenever V_(PWM) _(_) _(Q1) and V_(PWM) _(_) _(Q3) are high, i.e., corresponding to a positive voltage V_(AB) input to the transformer 120, and negative whenever V_(PWM) _(_) _(Q2) and V_(PWM) _(_) _(Q4) are high, i.e., corresponding to a negative voltage V_(AB) input to the transformer 120. Such a flux polarity indication B_(POL) could be latched whenever there is a change in the PWM waveforms, and this indication may be provided by the PWM generator 680 to the flux controller 670 so that the flux controller 670 is aware of the flux polarity. In many embodiments including, e.g., where B_(SAT) _(_) _(LO)=−B_(SAT) _(_) _(HI), it may not be necessary for the flux controller 670 to be aware of the flux polarity; the flux controller 670 could merely toggle between two polarities that it maintains.

In the following, sub-embodiments analogous to those described previously regarding the first embodiment will be described. Additional detail regarding the flux controller 670 and PWM generator 680 are provided in FIGS. 9 and 10, including techniques for balancing the magnetic flux. Note that this additional detail and the techniques described below are largely applicable to the first two embodiment also, but are described in this third embodiment as it is considered the preferred embodiment.

FIG. 7 illustrates the magnetic flux B in the transformer core 126 over three cycles of the voltage converter 600, as well as an estimation of the magnetic flux as tracked in the controller 660. The waveforms 700 of FIG. 7 are analogous to those of FIG. 3, but, for ease of illustration, the PWM waveforms are omitted in FIG. 7.

In a sub-embodiment of a voltage converter 600, it is presumed that the input source voltage V_(IN) is constant and, therefore, the magnetic flux B may be estimated using a counter with a fixed increment/decrement. A waveform 730 corresponding to a voltage V_(AB) output by the power stage 110 and input to the transformer 120 is illustrated over 3 cycles of the voltage converter 600. A load step caused by, e.g., an increased power requirement of the load 150 causes the increasing pulse durations illustrated. This leads to an increased magnitude of the magnetic flux B within the transformer core 126, as illustrated in the magnetic flux B waveform 740.

A secondary-side voltage V_(CD) (not shown for ease of illustration) is rectified leading to a rectified voltage V_(rect) having a waveform 760 as illustrated in FIG. 7. Note that the rectified voltage V_(rect) is slightly delayed relative to the transformer 120 input voltage V_(AB). The rectified voltage V_(rect) is input to the flux controller 670 where it is compared against a threshold V_(rect) _(_) _(thresh), e.g., using a comparator circuit, to yield the binary output V_(rect) _(_) _(comp), as illustrated in the waveform 770. The threshold V_(rect) _(_) _(thresh) is chosen to be at some value between 0 and an expected value of V_(rect) when this voltage is high.

A counter within the flux controller 670 increments when V_(rect) _(_) _(comp) is high and the flux polarity B_(POL) is positive, and decrements when V_(rect) _(_) _(comp) is high and the flux polarity B_(POL) is negative. The resultant Count is illustrated in the waveform 750, and serves to provide a first-order estimation of the magnetic flux 740. The flux controller 670 monitors the Count and, if it extends outside of the range between Count_(LIM) _(_) _(LO) and Count_(LIM) _(_) _(HI), a high-flux condition is detected. In response to such detection, the flux controller 670 indicates to the PWM generator 680 that any ongoing PWM pulses should be truncated so that power being input to the transformer 120 is curtailed. An example of this is shown in FIG. 7, wherein the Count waveform 750 exceeds the count limit Count_(LIM) _(_) _(HI) at a time instant 751, which is detected by the flux controller 670. The flux controller 670 indicates to the PWM generator 680 that any ongoing PWM pulses must be disabled immediately. Shortly thereafter, PWM waveforms (not shown for ease of illustration), such as V_(PWM) _(_) _(Q1) and V_(PWM) _(_) _(Q3) that control power switches Q₁, Q₃ within the power stage 110, are set low. This, in turn, shortens the positive pulse 735 of the transformer input voltage V_(AB) during cycle 3, thereby stopping additional magnetic flux B from being induced into the transformer core 126. Provided the safety margin Δ is adequate, the described technique prevents the magnetic flux B from exceeding the saturation limit B_(SAT) _(_) _(HI). This is shown in the magnetic flux B waveform 740.

In a further sub-embodiment, there is no presumption that the input voltage V_(IN) is constant, and the value of the rectified voltage V_(rect) is used to account for the variation in the input voltage V_(IN) and its effect on the magnetic flux B. Such an embodiment is analogous to that described for the first embodiment in conjunction with FIG. 4, with the primary difference being that the rectified voltage V_(rect) must be assigned an appropriate polarity before being added to the Count. Such a Count may be given by:

$\begin{matrix} {{{Count} = {{\Delta \; {BN}_{2}A} = {T*{\sum\limits_{k_{0}}^{k_{0} + K}{{v_{rect}(k)}*{B_{{POL}\;}(k)}}}}}},{{{{over}\mspace{14mu} {the}\mspace{14mu} {period}\mspace{14mu} {from}\mspace{14mu} k_{0}\mspace{14mu} {to}\mspace{14mu} k_{0}} + {{K.{wherein}}\mspace{14mu} {B_{POL}(k)}}} = \left\{ \begin{matrix} {{{+ 1}\mspace{14mu} {for}\mspace{14mu} {flux}\mspace{14mu} {increases}},} \\ {{{- 1}\mspace{14mu} {for}\mspace{14mu} {flux}\mspace{14mu} {decreases}},} \end{matrix} \right.}} & (10) \end{matrix}$

N₂ is the number of turns in a secondary winding 124 a, 124 b and

A is the cross-sectional area of the transformer 120.

Note that the flux polarity B_(POL) does not change within each pulse of the rectified voltage V_(rect), and that the flux polarity B_(POL) alternates from one pulse of the rectified voltage V_(rect) to the next.

FIG. 8 illustrates waveforms 800 corresponding to the further sub-embodiment of the third embodiment. The voltage V_(VB) provided to the transformer 120 has a step increase 831 in its value during a positive flux polarity of cycle 2, as shown in the V_(AB) waveform 830. This causes an increase in the rate 841 at which the magnetic flux B is increasing as shown in the flux waveform 840, and also causes a step increase 871 in the rectified voltage V_(rect), as shown in its waveform 870. The flux estimation 850 based upon a Count as given by equation (10) tracks 851 this increased magnetic flux B rate. The Count does not reach the upper count limit Count_(LIM) _(_) _(HI), during cycle 2. However, the increased magnitude of the voltage V_(rect) causes the improved count to drop below the lower count limit Count_(LIM) _(_) _(LO) at time t=t_(EXC) during the negative flux polarity of cycle 2. Detection that the flux estimation (Count) reaches a count limit Count_(LIM) _(_) _(LO), Count_(LIM) _(_) _(HI) causes the flux controller 670 to provide an indication to the PWM generator 680 that any ongoing PWM pulse should be truncated. This results in the negative V_(AB) pulse 833 and the negative-flux rectified voltage V_(rect) pulse 873 during cycle 2 being shortened relative to the pulses that would be generated if no high-flux condition were detected. While the flux estimation given by Count falls below the lower limit Count_(LIM) _(_) _(LO), the magnetic flux B of the transformer core 126 stays bounded within the flux limits B_(SAT) _(_) _(HI), B_(SAT) _(_) _(LO), i.e., the transformer core 126 does not reach a flux saturation level.

FIG. 9 illustrates a portion of a controller 960 such as that used in the voltage controller of the three embodiments described previously. In addition to limiting the magnetic flux B, the controller 960 also balances the positive and negative flux excursions in order to drive the long-term average flux to zero. The controller 960 of FIG. 9 includes a flux controller 970, a PWM generator 980, and a duty cycle determiner 990. The controller 960 of FIG. 9 may be implemented using electrical circuitry including processors and memory, as similarly explained regarding the controller 160 of FIG. 1. For ease of explanation, the controller 960 will be described as being part of the voltage converter 600 of FIG. 6, but it should be understood that the techniques implemented within the controller 960 could similarly be incorporated into the voltage converters 100, 500 of FIGS. 1 and 5.

The duty cycle determiner 990, which may be part of the PWM generator 980 in some implementations, uses the output load voltage V_(O) to determine a duty cycle (d) for the PWM generator 980. In a typical implementation, the output load voltage V_(O) is compared against a target voltage V_(TARGET) to generate an error voltage V_(ERR) (not shown). This error voltage V_(ERR) then feeds a duty cycle controller, such as a proportional-integral-derivative (PID) controller (not shown for ease of illustration), which determines whether the duty cycle (d) should be increased or decreased and by how much. Because the operation of PID controllers is well-known in the art, such conventional operation are not described further herein. The resultant duty cycle (d) is typically updated once per switching cycle of the voltage converter 600, and provided to the PWM generator 980. Note that the target voltage V_(TARGET) is typically stored within a memory of the controller 960, and may be set during a configuration or calibration of the voltage converter 600.

The flux controller 970 includes a flux estimator 972, a flux balancer 974, and a flux limiter 976. The flux estimator 972 inputs one or more of an input voltage V_(AB) from the primary side of a voltage converter, a voltage V_(CD) across the secondary winding of a voltage converter, and a rectified voltage V_(rect) on the secondary side of a voltage converter. A flux polarity B_(POL) may also be provided to the flux estimator 972, e.g., from the PWM generator 980, in some implementations, e.g., those in which the rectified voltage V_(rect) is used for estimating magnetic flux B. The flux estimator 972 estimates the magnetic flux B within the transformer core 126 based upon the input voltage. The flux estimate B_(EST) may be determined based upon a Count having a fixed increment/decrement, or on a Count having increment/decrement values determined by the input voltage. Such techniques for estimating the flux B are as described in the voltage converters 100, 500, 600 of FIGS. 1, 5, and 6. The estimated flux B_(EST) is provided to the flux balancer 974 and the flux limiter 976.

The flux limiter 976 uses the flux estimate B_(EST) (e.g., Count) to detect a high-flux condition. Such detection techniques are described above for the voltage converters 100, 500, 600 of FIGS. 1, 5, and 6, and, hence, such techniques will only be briefly summarized here.

Flux limits B_(LIM) _(_) _(HI), B_(LIM) _(_) _(LO) are provided to or stored within the flux limiter 976. These limits B_(LIM) _(_) _(HI), B_(LIM) _(_) _(LO) may be stored within a memory of the flux limiter 976, or within a memory otherwise located within the controller 960. As explained regarding the voltage converters 100, 500, 600 of FIGS. 1, 5, and 6, count limits Count_(LIM) _(_) _(HI), Count_(LIM) _(_) _(LO), which are examples of B_(LIM) _(_) _(HI), B_(LIM) _(_) _(LO), are determined based upon parameters such as a flux saturation limit B_(SAT) of a transformer core, the turns (e.g., N1, N2) within windings of a transformer, and a safety margin Δ. Typically, the limits B_(LIM) _(_) _(HI), B_(LIM) _(_) _(LO) have the same magnitude, but are of opposite polarity.

The flux limiter 976 monitors the flux estimate B_(EST) (e.g., Count) and constantly compares it against the flux limits B_(LIM) _(_) _(HI), B_(LIM) _(_) _(LO) (e.g., Count_(LIM) _(_) _(HI), Count_(LIM) _(_) _(LO)). If the flux estimate B_(EST) falls outside of the range {B_(LIM) _(_) _(HI), B_(LIM) _(_) _(LO)}) indicated by the flux limits, the flux limiter 976 provides an indication C that any active PWM pulse needs to be immediately truncated (clamped), so as to disable all power switches and, in turn, curtail any power from being input to the transformer 120. Note that while the flux limiter 976 serves to protect against flux saturation in the transformer 120, the described clamping of the PWM waveforms reduces the power being supplied to the load 150 of the voltage converter 600, and may serve to create a non-zero bias in the average flux within the transformer core 126. These problems may be at least partially mitigated by actively balancing the positive and negative flux excursions.

The flux balancer 974 uses the provided flux estimate BEST to generate a duty cycle adjustment Δd_(POS) that is used to remove any bias in the long-term magnetic flux, i.e., to drive the average flux to zero. In an exemplary technique, the flux balancer 974 latches a peak positive value B_(MAX) _(_) _(EST) of the flux estimate B_(EST) and a peak negative value B_(MIN) _(_) _(EST) of the flux estimate B_(EST) for each cycle of the voltage converter 600. This may be accomplished by monitoring the flux estimate B_(EST) and storing these peaks, or the peak values B_(MAX) _(_) _(EST), B_(MIN) _(_) _(EST) may be latched using edges of a voltage V_(AB), V_(CD), V_(rect) or using edges of the PWM waveforms, e.g., V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2). A difference in the peak values is generated for each switching cycle, e.g., ΔB=B_(MAX) _(_) _(EST)−B_(MIN) _(_) _(EST). This difference ΔB is integrated or low-pass filtered over several switching cycles to generate a filtered difference ΔB_(FILT). The filtered difference ΔB_(FILT) is then used to generate a duty cycle adjustment Δd_(POS), which is provided to the PWM generator 980. If the filtered difference ΔB_(FILT) is zero, then the flux is perfectly balanced between positive and negative half cycles, and the duty cycle adjustment Δd_(POS) may be left at zero. If the filtered difference ΔB_(FILT) is positive, this indicates a positive flux bias that needs to be compensated by reducing the time interval when positive voltage is applied across the input V_(AB) to the transformer 120. This is accomplished by setting the positive duty cycle adjustment Δd_(POS) to a negative value, thereby reducing the duty cycle of the positive interval and, correspondingly, increasing the duty cycle of the negative interval. (Within a switching cycle, the net energy transfer and the average duty cycle is not changed by the balancing.) The amount of the duty cycle adjustment Δd_(POS) may be determined as a function of the filtered difference ΔB_(FILT), e.g., Δd_(POS)=f(ΔB_(FILT)), via table look-up or via a similar mapping technique.

The PWM generator 980 includes a core PWM generator 982, duty cycle adjustment summation circuits 984 a, 984 b, and PWM waveform truncation/clamping circuits 988 a, 988 b. The duty cycle adjustment summers 984 a, 984 b input the duty cycle d and the duty cycle adjustment Δd_(POS), and generate separate duty cycles d_(POS), d_(NEG) for the positive and negative intervals of a switching cycle. The average of the separate duty cycles d_(POS), d_(NEG) for a given switching cycle is the same as the duty cycle d, i.e., the duty cycle adjustment Δd_(POS) effectively shifts energy between the positive and negative intervals of a switching cycle, but does not change the overall energy provided during that switching cycle.

The core PWM generator 982 inputs the separate duty cycles d_(POS), d_(NEG) and uses these to generate PWM waveforms. The truncation circuits 988 a, 988 b input the PWM waveforms from the core PWM generator 982 and, if instructed by the flux limiter 976 signal C, clamp pulses within the PWM waveforms.

The controller 960 described above serves to prevent flux saturation within the transformer core 126 by implementing a fast-acting clamp of the PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q4) that are used for switching power to the transformer 120, and to balance the magnetic flux B by implementing a slow-acting balancing of the flux using a filtered flux estimate ΔB_(FILT). However, any clamping of the PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3), V_(PQM) _(_) _(Q4) will deny needed and expected power to the load 150 of the voltage converter 600, at least temporarily. In addition to the undesired consequence that the output voltage V_(O) will drop, the duty cycle determiner 990 (e.g., PID controller) will attempt to compensate for this voltage drop as if it were caused by a change in the load requirements. The net effect of these actions is that transients (including, potentially, oscillations) will be induced on the output voltage V_(O) when the PWM waveforms are clamped. In an improved controller, the clamping of a PWM pulse is also accompanied by a duty cycle adjustment to compensate for the clamped pulse, and, thereby, more immediately balance the flux between positive and negative excursions.

FIG. 10 illustrates a controller 1060 that is largely the same as the controller 960 of FIG. 9, and the common circuits therein will not be described below. In addition to generating a clamping indication signal C, the flux limiter 1076 also generates a duty cycle adjustment Δd_(POS) _(_) _(FAST). Rather than merely curtailing power from being input to the transformer 120 and/or waiting for the slow-acting flux balancer 974 to balance the positive and negative flux excursions, the duty cycle adjustment Δd_(POS) _(_) _(FAST) serves to more immediately compensate for a clamped PWM pulse. To provide an explicit example, consider a situation in which the positive PWM pulse interval within a cycle of the voltage converter 600 is reduced by 10% due to the clamping indication signal C. In conjunction with this, the flux limiter 1076 would also generate a duty cycle adjustment Δd_(POS) _(_) _(FAST) indicating that the negative PWM pulse interval within that cycle should be increased by 10%. By effectively shifting energy transfer from the positive to the negative interval, the overall energy transfer through the transformer 120 during the switching cycle is unaffected by the clamping. While this more immediate balancing reduces the burden of the (slow-acting) flux balancer 974, the flux balancer 974 is still necessary to correct imbalance caused by anomalies other than detection of a high-flux condition and clamping of the output PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q4). For example, load steps that are small enough to not cause high-flux conditions may still cause imbalance which should be corrected, and voltage bias on the transformer input may cause imbalance which should be corrected.

The PWM generator 1080 is modified such that it inputs and uses the fast-acting duty cycle adjustment Δd_(POS) _(_) _(FAST). As illustrated in FIG. 10, additional summation circuits 1086 a, 1086 b are used to adjust the positive and negative duty cycles d_(POS), d_(NEG). Other techniques for making this duty cycle adjustment are also possible. For example, the slow-acting duty cycle adjustment Δd_(POS) and the fast-acting duty cycle adjustment Δd_(POS) _(_) _(FAST) could be summed before being provided to the PWM generator 1080.

The above embodiments are described in the context of a full-bridge voltage converter in which the power input to a transformer is controlled by the duty cycles of PWM waveforms that control power switches. Of particular note, and as illustrated in the waveforms 300 of FIG. 3 which may be generated by the voltage converter 100 of FIG. 1, the PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q3) that enable power switches Q₁ and Q₃ are both high at the same time and both low at the same time. In fact, a single generated waveform could be used to control both of these power switches Q₁, Q₃. Likewise, the PWM waveforms V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q4) that enable power switches Q₂ and Q₄ are both high at the same time and both low at the same time. The power input to the transformer 120 is controlled by adapting the duty cycles of these waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q3), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q4). However, it should be recognized that other techniques for controlling the power input to the transformer 120 may also be used in conjunction with the flux estimation and overflux protection techniques described above. Such other techniques for controlling power input, e.g., phase-shifted control, have advantages such as zero-voltage switching (ZVS) in some applications.

FIG. 11 illustrates waveforms 1100 in which a type of phase shifting of the PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q4), V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3) is used to control the power input to the transformer 120. The PWM waveform 1110 a for V_(PWM) _(_) _(Q1), which controls power switch Q₁, has a nominally fixed duty cycle (e.g., 50%). The PWM waveform 1110 b for V_(PWM) _(_) _(Q4), which controls power switch Q₄, is an inverted version of the PWM waveform 1100 a for V_(PWM) _(_) _(Q1). Similarly, the PWM waveforms 1120 a, 1120 b for V_(PWM) _(_) _(Q2), V_(PWM) _(_) _(Q3) are inverted versions of each other. The PWM waveform 1120 a for V_(PWM) _(_) _(Q2) is nominally a delayed (phase shifted) version of the PWM waveform 1110 a for V_(PWM) _(_) _(Q1). The amount of the phase shift (delay) for a given cycle of the voltage converter determines the energy transfer to the transformer 120 during that cycle. The PWM waveforms 1100 show 3 cycles, each having a corresponding phase shift PS1, PS2, PS3, wherein the power transfer is increasing over time as the result of, e.g., an increased power requirement of the load 150. The PWM waveforms 1110 a, 1110 b, 1120 a, 1120 b lead to the transformer input voltage V_(AB), which has a waveform 1130 as illustrated in FIG. 11.

The waveforms 1130, 1140, 1150 for the voltage V_(AB), magnetic flux B, and flux estimate Count are largely the same as the waveforms 330, 340, 350 of FIG. 3. The flux estimate Count may be determined based upon the transformer input voltage V_(AB), the transformer secondary voltage V_(CD), or some other voltage, e.g., V_(rect), in the conditioning circuit 140, as described in the prior embodiments. At time t=t_(EXC), the flux controller 170, 570, 670 detects that the flux estimate Count has exceeded a flux limit Count_(LIM) _(_) _(HI). The flux controller 170, 570, 670 indicates this high-flux condition 1151 to the PWM generator 180, 580, 680 which, in response, truncates the pulse 1123 b that starts in cycle 2 of the PWM waveform 1120 a for V_(PWM) _(_) _(Q3). Because the PWM waveform 1120 a for V_(PWM) _(_) _(Q3) is an inverted version of the PWM waveform 1120 a for V_(PWM) _(_) _(Q3), the rising edge of the V_(PWM) _(_) _(Q3) pulse 1123 a during cycle 3 is advanced in conjunction with this truncation. Stated alternatively, the phase shift PS3 that would normally be generated for the PWM waveforms 1120 a, 1120 b for V_(PWM) _(_) _(Q2) V_(PWM) _(_) _(Q3) during cycle 3 is modified to yield the reduced phase shift PS3 _(mod). The modified phase shift PS3 _(mod) (truncated PWM pulses), in turn, causes a truncation of the voltage pulse 1133 supplied to the transformer input V_(AB). Because this pulse 1133 is shortened, energy transfer to the transformer 120 is curtailed, and the magnetic flux density B of the transformer core 126 stays bounded within the saturation limits B_(SAT) _(_) _(HI), B_(SAT) _(_) _(LO). (Note that small delays are incurred between detecting the high flux condition, truncating the PWM pulse 1113 a, and truncating the V_(AB) pulse. For ease of illustration, these delays are not shown.)

As described above and illustrated in FIG. 11, the PWM waveforms 1120 a, 1120 b for V_(PWM) _(_) _(Q2) V_(PWM) _(_) _(Q3) are modified to limit the transformer flux B. Alternatively, the PWM waveforms 1110 a, 1110 b for V_(PWM) _(_) _(Q1) V_(PWM) _(_) _(Q4) could be modified. Such an alternative is not preferred in most applications, as typical phase-shift control already alters the PWM waveforms 1120 a, 1120 b for V_(PWM) _(_) _(Q2) V_(PWM) _(_) _(Q3) for controlling the power to a load 150. Requiring modification of the PWM waveforms 1110 a, 1110 b for V_(PWM) _(_) _(Q1) V_(PWM) _(_) _(Q4) may not be feasible in such applications.

Note that the flux balancing techniques described in conjunction with FIGS. 9 and 10 are also applicable to voltage converters using phase-shift control, by mapping the phase shifts (e.g., PS1, PS2, PS3) into duty cycles and slow-acting duty cycle adjustments (e.g., Δd_(POS)), and phase shift modifications (e.g., PS3-PS3 _(mod)) into fast-acting duty cycle adjustments (e.g., Δd_(POS) _(_) _(FAST)).

The above embodiments have been described in the context of a full-bridge voltage converter. However, the overflux protection and flux balancing techniques described above are also applicable to other isolated topologies. The incorporation of these techniques into an active clamp forward (ACF) voltage converter are described next. Note that these techniques make use of a rectified voltage V_(rect), in much the same manner as the full-bridge voltage converter 600 of FIG. 6. Only those aspects of the ACF voltage converter that are markedly different from that of the full-bridge converter 600 are described below. Also note that ACF voltage converters are well known in the art, and, hence, their conventional operation is not described in detail.

The ACF voltage converter 1200 of FIG. 12 includes a power stage 1210, a transformer 1220, an isolator 1230, a conditioning circuit 1240, and a controller 1260. An input power source V_(IN) provides power to the voltage converter 1200, and the voltage converter 1200 supplies output power to a load 1250.

The power stage 1210 includes power switches Q₁, Q₂, and a driver stage 1212 for driving the power switches Q₁, Q₂. The power switches Q₁, Q₂, are controlled to provide power to the transformer 1220. The transformer 1220 is modelled as having a leakage inductance L_(lk) and a magnetizing inductance L_(mag). The transformer 1220 includes a primary winding 1222 having N₁ turns, a secondary winding 1224 having N₂ turns, and a core 1226. The isolator 1230 buffers PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2) that are generated by the controller 1260 and that control the power switches Q₁, Q₂ within the power stage 1210. The conditioning circuit 1240 rectifies the voltage provided on the secondary side of the transformer 1220 using power switches Q_(SR1) and Q_(SR1). The conditioning circuit 1240 also filters the rectified voltage V_(rect) using inductor L_(O) and capacitor C_(O), and provides a filtered voltage V_(O) to the load 1250. The controller 1260 provides control signals to the power switches Q_(SR1) and Q_(SR1) for the voltage rectification, and the PWM generator 1280 therein generates the PWM waveforms V_(PWM) _(_) _(Q1), V_(PWM) _(_) _(Q2). The controller 1260 also includes a flux controller 1270 that detects high-flux conditions and, in conjunction with the PWM generator 1280, limits the flux being input to the transformer 1220.

The flux controller 1270 is similar to the flux controller 670 of FIG. 6. However, the measured rectified voltage V_(rect) of FIG. 12 is not sufficient for flux estimation. The flux controller 1270 also measures a voltage corresponding to the drain-source voltage V_(ds) across the rectification power switch Q_(SR1). (The rectified voltage V_(rect) and/or the drain-source voltage V_(ds) may need to be shifted, e.g., using a resistor divider, before being input to the controller 1260. For ease of illustration, this is not shown.) The flux estimation is then based upon the difference between the rectified voltage V_(rect) and the drain-source voltage V_(ds). This voltage difference corresponds to the voltage V_(CD) across the secondary winding 1224 of the transformer 1220. The flux controller 1260 uses the voltage difference (corresponding to the voltage V_(CD)) to estimate the magnetic flux using techniques as described regarding the flux controller 670 of FIG. 6. The estimated magnetic flux is then used to detect high-flux conditions and, responsive to such detection, to modify the PWM waveforms generated by PWM generator 1280 in order to prevent flux saturation in the transformer core 1226.

FIG. 13 illustrates a method 1300 for avoiding magnetic flux saturation within a transformer of a voltage converter. This method may be implemented, e.g., within a controller of the voltage converter. The techniques of this method 1300 are similar to those described above regarding the voltage converters 100, 500, 600, 1100, 1200 of FIGS. 1, 5, 6, 11 and 12.

In a first step 1310, PWM waveforms are generated for controlling one or more power switches within the voltage converter. Each of these PWM waveforms is comprised of a series of PWM pulses, wherein at least one of the duty cycle, switching frequency, and phase shifting of the PWM waveforms determines the amount of power transferred to the transformer. The magnetic flux within the transformer is estimated 1320 based upon a voltage across the primary winding of the transformer and/or a voltage within a conditioning circuit coupled to the secondary side of the transformer, in order to generate a magnetic flux estimate B_(EST). The magnitude of the flux estimate BEST is compared 1330 against a flux limit B_(LIM) to determine if a saturation flux level is being approached. If the magnitude of the flux estimate B_(EST) exceeds the flux limit B_(LIM), corrective actions are taken to curtail power from being provided to the transformer. More particularly, any ongoing PWM pulse(s) within the PWM waveforms is (are) truncated 1335 in this situation. After the PWM pulse truncation 1335 or if no truncation is needed, the PWM waveforms are provided 1340 to the power switches in order to control the power being provided to the transformer.

As used herein, the terms “having”, “containing”, “including”, “comprising” and the like are open-ended terms that indicate the presence of stated elements or features, but do not preclude additional elements or features. The articles “a”, “an” and “the” are intended to include the plural as well as the singular, unless the context clearly indicates otherwise.

It is to be understood that the features of the various embodiments described herein may be combined with each other, unless specifically noted otherwise.

Although specific embodiments have been illustrated and described herein, it will be appreciated by those of ordinary skill in the art that a variety of alternate and/or equivalent implementations may be substituted for the specific embodiments shown and described without departing from the scope of the present invention. This application is intended to cover any adaptations or variations of the specific embodiments discussed herein. Therefore, it is intended that this invention be limited only by the claims and the equivalents thereof. 

1-20. (canceled)
 21. A voltage converter, comprising: a power stage comprising one or more power switches; a conditioning circuit operable to supply power to a load of the voltage converter; a transformer configured to couple the power stage to the conditioning circuit; and a controller operable to: estimate magnetic flux within the transformer based upon a voltage measured within the voltage converter; and generate control signals that drive the one or more power switches based upon the estimated magnetic flux.
 22. The voltage converter of claim 21, wherein the controller is further operable to generate the control signals so as to balance the estimated magnetic flux such that any positive or negative bias in the estimated magnetic flux is reduced.
 23. The voltage converter of claim 22, wherein the generated control signals are pulse-width-modulated (PWM) waveforms comprised of a sequence of switching cycles, wherein each switching cycle comprises a positive pulse and a negative pulse; and wherein balancing the estimated magnetic flux is performed by increasing a duration of one of the positive and negative pulses, and decreasing a duration of the other of the positive and negative pulses, such that the sum of the durations for the positive and negative pulses remains substantially unchanged.
 24. The voltage converter of claim 21, wherein the controller is further operable to: detect an overflux condition in which a magnitude of the estimated magnetic flux has exceeded a flux magnitude limit for the transformer; and responsive to detecting the overflux condition, alter the generated control signals so as to curtail power transfer from the power stage to the transformer.
 25. The voltage converter of claim 21, wherein the controller is further operable to: detect an overflux condition in which a magnitude of the estimated magnetic flux has exceeded a flux magnitude limit for the transformer; responsive to detecting the overflux condition, alter the generated control signals so as to curtail a current power transfer from the power stage to the transformer; and further alter the generated control signals so as to shift power between positive and negative half cycles, thereby compensating for the curtailed current power transfer.
 26. The voltage converter of claim 21, wherein the magnetic flux is estimated using a volt-second measure.
 27. The voltage converter of claim 26, wherein estimating the magnetic flux using the volt-second measure is performed by: periodically measuring the voltage within the voltage converter; and maintaining a running sum of the measured voltages.
 28. The voltage converter of claim 21, wherein the voltage measured within the voltage converter is a voltage across a primary winding of the transformer.
 29. The voltage converter of claim 21, wherein the voltage measured within the voltage converter is a voltage across a secondary winding of the transformer, or is a voltage within the conditioning circuit.
 30. A method within a voltage converter comprised of a power stage having one or more power switches, a conditioning circuit operable to supply power to a load of the voltage converter, and a transformer configured to couple the power stage to the conditioning circuit, the method comprising: estimating magnetic flux within the transformer based upon a voltage measured within the voltage converter; and generating control signals that drive the one or more power switches based upon the estimated magnetic flux.
 31. The method of claim 30, wherein the control signals are generated so as to balance the estimated magnetic flux such that any positive or negative bias in the estimated magnetic flux is reduced.
 32. The method of claim 31, wherein the generated control signals are pulse-width-modulated (PWM) waveforms comprised of a sequence of switching cycles, wherein each switching cycle comprises a positive pulse and a negative pulse; and wherein balancing the estimated magnetic flux is performed by increasing a duration of one of the positive and negative pulses, and decreasing a duration of the other of the positive and negative pulses, such that the sum of the durations for the positive and negative pulses remains substantially unchanged.
 33. The method of claim 30, further comprising: detecting an overflux condition in which a magnitude of the estimated magnetic flux has exceeded a flux magnitude limit for the transformer; and responsive to detecting the overflux condition, altering the generated control signals so as to curtail power transfer from the power stage to the transformer.
 34. The method of claim 30, further comprising: detecting an overflux condition in which a magnitude of the estimated magnetic flux has exceeded a flux magnitude limit for the transformer, responsive to detecting the overflux condition, altering the generated control signals so as to curtail a current power transfer from the power stage to the transformer; and further altering the generated control signals so as to shift power between positive and negative half cycles, thereby compensating for the curtailed current power transfer.
 35. The method of claim 30, wherein the magnetic flux is estimated using a volt-second measure.
 36. The method of claim 35, wherein estimating the magnetic flux using the volt-second measure is performed by: periodically measuring the voltage within the voltage converter and maintaining a running sum of the measured voltages.
 37. The voltage converter of claim 30, wherein the voltage measured within the voltage converter is a voltage across a primary winding of the transformer.
 38. The voltage converter of claim 30, wherein the voltage measured within the voltage converter is a voltage across a secondary winding of the transformer, or is a voltage within the conditioning circuit. 